Cavity Resonator For MR Systems

ABSTRACT

A magnetic resonance apparatus in embodiments of the invention may include one or more of the following features: (a) a coil having at least two sections, (b) the at least two sections having a resonant circuit, (c) the at least two sections being wirelessly coupled or decoupled, (d) the at least two sections being separable, (e) several openings allowing a subject to see and be accessed through the coil, (f) at least one cushioned head restraint, and (g) a subject input/output device providing visual data from in front and behind of the coil respectively; wherein the input/output device is selected from the group consisting of mirrors, prisms, video monitors, LCD devices, and optical motion trackers.

CROSS REFERENCE

This application is a divisional application from U.S. application Ser. No. 10/440,641, filed May 19, 2003, now pending, which claims benefit of Provisional Application Ser. No. 60/381,356, filed May 17, 2002, the contents of which are incorporated herein by reference in their respective entireties.

FIELD OF THE INVENTION

The present invention relates to a cavity resonator coil for use in magnetic resonance systems.

BACKGROUND OF THE INVENTION

There are many previously known resonators for use in magnetic resonance (MR) systems for imaging and spectroscopy. For example, one previously known device is commonly known as a birdcage resonator. These previously known birdcage resonators typically comprise a plurality of circumferentially spaced inductive/capacitive elements connected by inductive/capacitive end ring elements, which are driven at resonance by a Larmor radio frequency useful for nuclear magnetic resonance (NMR) systems. The object to be analyzed, e.g. the brain, is positioned within the resonator during the operation of the MR system.

One disadvantage of these previously known resonators, however, is that they typically use lumped element circuits (with discrete inductors and capacitors) to achieve resonance at the selected radio frequency. Because lumped element circuits lose more energy to radiation at high frequencies where the circuit is greater than 1/10 wavelength, the lumped element resonator is less efficient for high field MR imaging applications compared to lower field strengths. Because lumped element circuits are more radiative, they are electrically less efficient and have a lower Q factor. Similarly because conventional lumped element circuits such as the birdcage are more inductive, they resonate at lower frequencies than do the less inductive transmission line (TEM) circuits.

These previously known resonators, which use lumped element circuits, suffer from several additional disadvantages. One such disadvantage is non-uniform current distributions which result in decreased homogeneity, decreased fill factor, and increased electric field losses. Especially at higher frequencies and for larger (clinical) volumes, lumped element resonators may achieve self-resonance below the desired frequency of operation as well as increased electromagnetic radiation losses.

A distributed circuit, cavity resonator for NMR systems disclosed by Vaughan in U.S. Pat. No. 5,744,957 overcomes the above-mentioned disadvantages of the previously known devices. Vaughan discloses a cavity resonator having coaxial inner and outer cylindrical walls separated by a dielectric region. Spaced conductive end walls extend across the inner and outer walls at each axial end of the coil so that the inner, outer, and end walls together form an approximate cavity. The inner, outer, and end walls can, for example, be coated with a thin foil conductive material, such as copper, silver, or gold. In doing so, the coil imitates a coaxial line segment made resonant at Larmor frequencies useful for MR, such as 64 MHz (1.5 T), 175 MHz (4.1 T) or 170 MHz (4 T).

The apparatus disclosed by Vaughan provides a cavity resonator coil overcoming the problems of conventional coils discussed above, providing for a substantial improvement in signal to noise ratio (SNR). The coil will also resonate and operate efficiently at higher Larmor frequencies for the higher static magnetic now available at 3 T and above. Because the SNR from MR samples increases with the magnet field strength, the ability of this coil to resonate and operate efficiently at higher frequencies means that it can be used at high field strengths to obtain further SNR gains. This increase in signal to noise ratio provides a substantially improved image of the object to be analyzed within the resonator during the operation of the MR system, for example.

The resonator disclosed by Vaughan has proven effective in MR systems providing increased SNR, homogeneity, transmit efficiency, fill factor, decreased electric field losses, and higher operational frequencies. However, there are still some problems associated with both the resonator disclosed by Vaughan and the previously known lumped element resonators.

An ideal clinical head coil for example would lend itself to the easiest and most comfortable subject positioning, leave the subject's face uncovered once the subject is in position, and would include these access and comfort features without compromising coil performance, safety and reliability. It is preferable for a head coil to be both comfortable and accessible for the subject and easy to use for the technician. However, it is difficult to provide comfort and accessibility for the subject and ease of use for the technician and maintain a high coil performance. The ideal coil should have a removable top as well, to allow for comfortable subject positioning in the coil. Furthermore, some commercial systems don't provide the space for a coil that slides over a subject's head. Accordingly, several commercial coil designs already incorporate this “pop top” feature. However, these commercial coils that separate into halves are not popular with some research applications such as fMR. Apparently the electrical contacts that are broken and remade to open and close the coil each time a new subject is loaded, become unstable over time due to wear and oxidation, resulting in noise “spikes” and temporal instabilities often seen in EPI images for example. These electrical contacts are required to complete the end ring current paths in birdcages and similar coil structures. While commercial coils must meet rigorous FDA safety criteria, it could be imagined that electrical contacts in a coil might possibly pose safety risks in certain situations, especially where electrolytic bodily fluids were present.

Similarly, an ideal body coil might be as small as possible and fit close enough to the human trunk for efficient transmission to and reception from a region of interest, but allow room for subject comfort and access. The present body coils are built very large to allow for access and comfort, but as a consequence are very inefficient and are poorly couplet the MR region of interest in a body. RF power amplifiers of 35 kW and more are required to compensate for the inefficiencies of a body coil used in a 3 T magnet for example. Still, these coils provide little shoulder room for the largest human subjects.

Limb coils, especially leg coils, are similarly limited by conventional practice. A leg volume coil for example must be oversized to make room for a leg with a foot to be threaded through the cylindrical structure. Or a leg coil has a removable top to provide easier access for a closer fitting, more efficient coil. This latter coil however by conventional designs requires the problematic electrical contacts described for the head coil above.

Typical existing head-only MR systems are one-piece units. A significant problem with this structure is that many medical subjects do not possess the physical ability to manipulate their heads and bodies into the positions required for the MR without significant difficultly or pain. Typically, the subject must try and navigate their head into the small diameter of the head only system. This can be painful or impossible for most medical subjects who are asked to do this while lying on their back.

Because of the inherently low SNR of the MR signal, these signals must be acquired and averaged a sufficient number of times to improve the SNR to a significant value. MR data acquisition by signal averaging is highly intolerant of motion in the MR sample or subject. Accordingly, human subjects are required to remain motionless for the duration of an MR scan, sometimes lasting 30 minutes or more. Movement will result in lower resolution images and in image “ghosting”, thereby limiting the diagnostic quality of an image and often requiring a repeated imaging session. To minimize head motion for example, MR operators will often insert padding around the subject's head to provide head restraint. While this has the effect of reducing the subject's head movement, it does not eliminate all of the subject's head movement. Further, all of the padding placed around the subject's head can apply uncomfortable pressure and can intensify the subject's feelings of claustrophobia. Therefore, the purpose behind having a high performance coil with a better signal to noise ratio is defeated if the subject cannot remain still.

Another problem associated with many MR protocols, is they can be painfully loud. Typically, subjects are given earplugs or headphones to muffle the noise (in most MR centers the subject can even bring their own cassette or CD to listen to). The acoustic noise is attributed to the electro motive forces generated by switched electrical currents in the wires of the magnet's gradient coils. Stronger magnet fields and stronger or faster gradient current switching generate greater acoustic amplitudes. While the methods mentioned above are generally effective for gradient noise reduction, coils must be built to larger and less efficient dimensions to accommodate the head restraint and hearing protection devices placed about the head.

Visual input/output is often required for a subject receiving an MR exam, for diagnostics or research. These I/O visual devices help to minimize claustrophobia, provide visual cues, and relay information from the MR operator. Visual I/O devices are typically mirrors, prisms, or active displays located above the subject's eyes. A problem with existing systems of this sort is that 1) they are often fixed in position which requires that a subject be adjusted to the device, and 2) they typically protrude above the head coil so as to preclude their use in close fitting head only MR systems, and in head gradient inserts used in whole body MR systems.

It has been shown that back planes on RF coils can function as an RF mirror to extend the uniformity of the coil's transverse RF magnetic field along the rotational or “z” axis of the coil. A back plane, also known as an end cap, can be used in a coil to make a shorter, and therefore more ergonomic, better shielded, and more electrically efficient coil for a desired field of view. Conventional cylindrical birdcage head coil, as mentioned above, typically do not have a back plane. The lack of a back plane together with the inherently shorter axial field of a birdcage require the birdcage head coil to be longer typically covering the subject's mouth and chin. This increased length of the birdcage has many problems. It creates a head coil, which can increase feelings of claustrophobia for the subject. Once inside of the head coil the subject's mouth is located immediately in front of the inside coil wall. A subjects breath pushed back into their face by the inside coil wall creates a very uncomfortable/claustrophobic feeling for the subject. This is an undesirable result since the MR exam may take 20 to 90 minutes. Additionally, general medical access and vocal communications are impeded with the coil extending over the subject's mouth and chin. Further, if the subject has a large head, nose, and/or chin it becomes increasingly difficult to fit the subject's head inside of the coil. Another additional disadvantage for coils not having end caps is additional electromagnetic energy is lost from the top of the coil and thus the coil is less efficient at high frequencies.

While a back wall in a head coil is more desirable for coil performance and ergonomics in relation to the subject's mouth and chin (i.e., with a back wall the head coil body can be shorter and thus the head coil does not have to extend over the chin), a back wall is undesirable for a couple of reasons. First, a back plane closes off one end of the coil giving the appearance of putting ones head into a bucket rather than an open cylinder. This can increase a feeling of claustrophobia for the subject. Second, the back plane limits access to the subject from the back of the magnet. In coils without back planes, leads for physiological monitors, anesthesia and/or respiratory hoses, EEG leads, communications lines, etc., can be passed. In these systems visual signal projection is often performed from the rear of a magnet and through the back of a coil to mirror or prism systems mounted above the subjects' eyes. Therefore, presently, head coil manufacturers must choose between the benefits of having a coil back plane or end cap or the benefits associated with access to the subject provided by head coils with no end cap.

As stated above, a problem associated with head coils is the amount of space provided inside of the coil. RF coils transmit MR stimulus to the subject and receive signals back most efficiently when the coil is as close as possible to the subject. Therefore, for RF coil performance considerations, space inside a coil should be only enough for subject comfort and for the inclusion of devices useful for safety, head stability, and communication with the subject. As stated above, normally a subject must wear earphones or plugs for hearing protection and have separate pads inserted around the head to hold the head motionless for the MR exam. Further, there is typically some sort of visual and/or audio communications device adjacent to the head so that the MR operator can communicate with the subject. However, the padding, hearing protection and communication equipment can not only make the MR experience uncomfortable for the subject but this equipment also occupies limited space within the head coil.

All of these problems listed above, individually and collectively, degrade the overall quality of NMR images and spectra, add to the discomfort of the subject, and limit subject access for the physician or researcher. Therefore, what is clearly needed is a high performance apparatus, which provides for increased signal to noise ratios and improved MR image quality, while overcoming the problems discussed above.

SUMMARY OF THE INVENTION

An magnetic resonance apparatus in embodiments of the invention may include one or more of the following features: (a) a coil having at least two sections, (b) the at least two sections having a resonant circuit, (c) the at least two sections being wirelessly coupled or decoupled, (d) the at least two sections being separable, (e) several openings allowing a subject to see and be accessed through the coil, (f) at least one cushioned head restraint, and (g) a subject input/output device providing visual data from in front and behind of the coil respectively; wherein the input/output device is selected from the group consisting of mirrors, prisms, video monitors, LCD devices, and optical motion trackers.

A magnetic resonance apparatus in embodiments of the invention may include one or more of the following features: (a) a coil having at least one head restraint, (b) a means for audio communication to a subject connected to the head restraint, (c) a means for active or passive protection for a subject's hearing, (d) at least three head restraints to provide a three-point head restraint, (e) a means to secure said head restraint to a subject's head, and (f) a head cushion.

A TEM coil providing MR imaging in embodiments of the invention may include one or more of the following features: (a) a coil providing at least two head restraints, (b) the head restraints having a means for audio communication to a subject, (c) a means for active or passive protection for a subject's hearing, (d) a head cushion to provide a three-point head restraint, (e) a means to secure said head restraints to a subject's head, and (f) a means to accept an audio signal input.

A magnetic resonance apparatus in embodiments of the invention may include one or more of the following features: (a) a coil having at least two separable sections, (b) an input/output device, (c) a track system located within an open face area in the coil, and (d) the input/output device being slideably mounted on said track.

A TEM coil in embodiments of the invention may include one or more of the following features: (a) an input/output device, (b) a track system located within an open face area in the coil, (c) the input/output device being slideably mounted on said track, and (d) the input/output device is selected from the group consisting of visual transducers, olfactory transducers, gustatory transducers, or auditory transducers to provide two way communication or stimulus.

An RF coil for magnetic resonance in embodiments of the invention may include one or more of the following features: (a) the coil comprising a plurality of sections, (b) the plurality of sections being with wireless connections and able to wirelessly couple electromagnetic energy between the plurality of sections or the plurality of sections being reactively decoupled, (c) the plurality of sections being separable, and (d) a guiding means to assure mutual alignment between said plurality of sections.

A method of manufacturing a magnetic resonance device in embodiments of the invention may include one or more of the following steps: (a) providing a coil having a plurality of sections; the plurality of sections being separable, (b) attaching a head restraint means to prevent movement of a subject's head, provide communication with the subject, and protect said subject's hearing, (c) inserting a slideable input/output device within an open window on said top section to provide subject with two way communication, (d) creating a rear projection slot providing a channel positioned in a back plane of said coil to provide access for a rear visual projection system.

A method of performing magnetic resonance imaging in embodiments of the invention may include one or more of the following steps: (a) providing a coil having a top section and a bottom section; said top section and bottom section being separable and wirelessly connected, (b) placing a subject within the bottom section, (c) placing the top section in electromagnetic communication with the bottom section, (d) providing a plurality of openings in the top section to allow a subject to see through said coil and be accessed through said coil, (e) providing at least one cushioned device for head restraint.

BRIEF DESCRIPTION OF THE DRAWINGS

FIG. 1 is an exploded view of a construction of a resonator.

FIG. 1 a is a profile view of a construction of a resonator according to FIG. 1.

FIG. 2 is an exploded view of an internal construction of a resonator according to an embodiment of the present invention.

FIG. 2 a is an exploded view of a resonator according to an embodiment of the present invention.

FIG. 2 b is a side profile diagram of a simulated subject's head within a resonator for the present invention.

FIG. 2 c is a profile view of a prior art bird cage coil.

FIG. 2 d is a profile view of a TEM cavity resonator.

FIG. 2 e is a profile view of a resonator according to an embodiment of the present invention.

FIG. 2 f is a profile view of a resonator according to an embodiment of the present invention.

FIG. 3 is an enlarged view of the exploded view of a resonator as shown in FIG. 2 a.

FIG. 4 is an exploded front profile of a resonator for the present invention.

FIG. 5 is a rear side profile view of a resonator for the present invention.

FIG. 6 is a front profile of a resonator for the present invention.

FIGS. 7 a, b, c, d compare lumped element resonant circuits to transmission line analogues.

FIGS. 8 a, b diagrammatically illustrate a coaxial cavity used for high frequency volume MR coils according to the invention.

FIGS. 9 a, b diagrammatically illustrate a tuned TEM resonator according to the invention.

FIG. 10 is a diagram of the modes of an eight element TEM resonator.

FIGS. 11 a, b, c, d, e show B₁ flux line representations for the five modes of an eight element TEM resonator, according to the invention.

FIG. 12 shows time dependent B₁ magnetic vector equipotentials for mode 1 of a head loaded coil according to the invention.

FIG. 13 is a sectional view of a portion of FIG. 12.

FIGS. 13 a, b show time-dependent B₁ contours for mode 1 of the phantom and head loaded resonator according to the invention.

FIGS. 14 a, b show alternative circuit models for a tuned TEM resonator according to the invention.

FIG. 15 is an elevation, in perspective, of a tuned TEM resonator for a high frequency, large volume MR coil, according to the invention.

FIG. 16 is a circuit diagram of a driven coaxial line element used in the present invention.

FIG. 17 is a diagram of transmission return loss showing resonances of a sixteen element resonator according to the invention.

FIG. 18 is an elevation, in perspective, of a dual frequency tunable TEM resonator for a high frequency, large volume MR coil, according to the invention.

FIG. 19 is a sectional view of a portion of FIG. 18.

DETAILED DESCRIPTION

To assist in an understanding of the invention, a preferred embodiment or embodiments will now be described in detail. Reference will be frequently taken to the figures, which are summarized above. Reference numerals will be used to indicate certain parts and locations in the figures. The same reference numerals will be used to indicate the same parts or locations throughout the figures unless otherwise indicated.

The present invention is not limited to only distributed circuit cavity resonator head coils, and may be employed in many of various types of MR head coil devices. It is to be further understood, moreover, the present invention may be employed in many of various types of MR devices and is not limited only to head coils. For purposes of illustration only, however, the present invention is below described in the context of cavity resonator head coils.

With respect to FIGS. 1 & 1 a, a general construction of a cavity resonator is shown. Additional structures and teachings for construction of a cavity resonator, which can be utilized in the present invention are discussed in U.S. Pat. No. 5,557,247, U.S. Pat. No. 5,744,957, U.S. Pat. No. 5,886,596, U.S. Provisional Application 60/135,269, U.S. Provisional Application 60/222,144, U.S. Provisional 60/378,111, and U.S. Provisional 60/373,808, which are herein incorporated by reference in their entirety. Generally a cavity resonator (coil) 10 is comprised of an electrical circuit tube/board 12, a front cavity wall component 14, a lateral cavity wall component 16, and a back cavity wall component 18 all contained within a coil shell 22.

With reference to FIG. 2, an exploded view of an internal construction of a resonator according to an embodiment of the present invention is shown. Generally coil 24 is comprised of electrical circuit tube/board 12 and 12′, front cavity walls 14 & 14′, lateral cavity walls 16 & 16′, and back cavity wall 18 & 18′ all contained within coil shell 22 & 22′. Electrical circuit tubes 12 and 12″ are generally comprised of circuit elements which may be transmission line elements including coaxial line, flat line, stripline, microstrip, wave guide or other distributed elements, inductors, capacitors, PIN diodes, or other lumped elements, printed or etched circuit boards, preamps, TR switches, phase shifters, amplitude modulators, and other electronics devices. Tubes 12 and 12′ are inductively coupled by mutual inductance of the current elements in each. Cavity walls 14,14′, lateral cavity walls 16,16′, and back cavity wall 18,18′ are all electromagnetic shields or conductive strips comprised of conductive foil to complete the circuit, to limit radiative losses and to provide a Faraday shield for the coil 24. Coil shells 22, 22′ are comprised of a nonconducting packaging material such as plastic or fiberglass to house the internal components of coil 24, which are discussed above. When combined, front wall 14′, tube 12′, lateral wall 16′, back wall 18′, and coil shell 22′ are combined to form top section 28. In addition, front wall 14, tube 12, lateral wall 16, back wall 18, and coil shell 22 are combined to form bottom section 26. The internal construction of coil 24 is only essential to the present invention to the extent that it agrees with the external construction as shown in FIGS. 2 a-6 and provides for some preferred manufacturing methods and materials. It is contemplated that coil 24 can have most any type of internal MR structure, however, preferably resonator 24 has a general internal structure similar to that of the teachings of U.S. Pat. No. 5,557,247, U.S. Pat. No. 5,744,957, U.S. Pat. No. 5,886,596, U.S. Provisional Application 60/135,269, U.S. Provisional Application 60/222,144, U.S. Provisional 60/378,111, or U.S. Provisional 60/373,808.

Through research it has been found that hospitals, physicians, and MR system operators prefer to have a coil, which comes apart in two halves for ease of subject accessibility. With respect to FIG. 2 a, an exploded view of an embodiment for a coil of the present invention is shown. In a preferred embodiment, coil 24 is comprised of a top section 28, and a bottom section 26. While FIGS. 2-6 show coil 24 having only a top 28 and bottom section 26, it is fully contemplated that coil 24 could have a plurality of sections without departing from the spirit of the invention. However, for the purposes of this discussion, coil 24 is characterized as having a top 28 and bottom section 26. Generally, since the two halves of coil 24 are wirelessly coupled through inductive or capacitive coupling, there is no need for electrical contacts to bind top section 28 with bottom section 26. Basically coil 24 is comprised of conductor elements located in top section 28 mutually coupled to elements in bottom section 26. This reactive coupling is possible utilizing structures similar to those in U.S. Pat. No. 5,557,247, U.S. Pat. No. 5,744,957, U.S. Pat. No. 5,886,596, U.S. Provisional Application 60/135,269, U.S. Provisional Application 60/222,144, U.S. Provisional 60/378,111, or U.S. Provisional 60/373,808. Coil 24 can be viewed as an array of resonant units (each unit comprised of a conductive element with cavity segment) all reactively coupled to each other. Thus there is no need for hard electrical contacts to transfer energy between top section 28 and bottom section 26, thus the energy is transferred wirelessly. Alternately, as shown in FIGS. 2 e and 2 f, a plurality of sections 112 are reactively decoupled and driven by independent transmitters, or received by independent receivers or both transmit and receive such as is used in parallel imaging. These separate resonant circuits not only make top section 28 and bottom section 26 separable from one another they also have the added benefit of preventing switched gradient current induced eddy currents in coil 24.

With reference to FIG. 2 c, previously known devices such as birdcage 100, discussed above, require electrical contacts to complete an end ring 102 circuit on each end. Birdcage coil 100 design has one or more end ring 102 circuits at each end of the coil design, which provide current return paths to separate legs that traverse between two rings 102. Thus, the operation of a birdcage coil 100 design relies on current flow through end rings 102. Therefore, separating birdcage 100 into two halves requires hard electrical contacts between the two halves to be broken. Electrical contacts provide many problems including being prone to wear, oxidation, intermittency, and potential safety hazards for the subject.

The current paths on conventional birdcage coils 100 are dependent on end rings 102 making birdcage 100 inductance dependent on the diameter of the coil. Large coils such as head and body coils are very inductive and therefore resonate at lower frequencies.

With reference to FIGS. 2 d, 2 e, and 2 f, resonant cavity 110 circuit of the present invention does not depend on a current return path on an end ring 102, as does a birdcage 100. The current return in the preferred embodiment occurs on its associated cavity wall 108 segment, creating an electrically shorter, and therefore less inductive, more current uniform, higher frequency, and more efficient circuit than an equal sized birdcage 100. The operational frequency of birdcage 100 is dependent on and limited by the inductive end ring 102. TEM or cavity resonator 110 whose operational frequency is not dependent on or limited by an end ring 102 however can obtain much higher frequencies.

The current paths on TEM resonator 110 are not dependent on end rings 102, but rather on cavity wall 108 to provide a “return” path for current elements 109. TEM coil 110 can therefore be arbitrarily large in diameter such as a large body coil, and still resonate at frequencies limited only by the size of an individual line element. Segmented TEM coils 110 shown in FIGS. 2 e and 2 f are shown to highlight the individual segments 108 or line elements 109 of which a TEM coil 110 is composed. Because the operation of TEM coil 110 does not depend on an end ring 102, segments 112 from coil 110 can be removed as shown without affecting the operational coil.

Therefore, the present invention utilizes top section 28 reactively coupled, inductively and/or capacitively, to bottom section 26 to allow for a separable design without the necessity of hard electrical contacts. The two sections of coil 24 are coupled reactively to one another so that all electrical circuits of coil 24 are sealed harmlessly inside dielectric coil packaging 27. The present invention not only makes coil 24 more accessible to subjects, it also minimizes or prevents any electrical shock hazard to the subject. Further, the separation of top section 28 and bottom section 26 assists in preventing eddy currents.

Another benefit of the reactive design of coil 24 is the ability to create an open window 29 substantially near the top of top section 28. As discussed above, a common problem with present systems is the coil giving the subject either an increased feeling of claustrophobia or not providing enough room for subjects with large heads, noses, and/or chins. Since, top section 28 has several openings 25, between inductively coupled elements of coil 24, the subject can freely see out of coil 24 and thus the feeling of claustrophobia is significantly reduced. Additionally, general medical access and vocal communications are not impeded due to open sections 29 & 25. Further, if the subject has a large head, nose, and/or chin, open window 29 allows the subject to fit comfortably within coil 24 as is depicted in FIG. 2 b. The use of open window 29 allows a larger head to fit, into a smaller, closer fitting, and therefore more efficient coil 24.

FIG. 3 shows an enlarged view of FIG. 2 a. With respect to FIG. 3, combination head restraints 30 and head cupped cushion 31 are shown. As stated above, regardless of the amount of padding used to prevent motion of the subject's head there is inevitably still some motion. Moreover, the padding can cause the subject some discomfort from compression and an increased feeling of claustrophobia. Combination head restraints 30 and head cushion 31 of the present invention not only provide an improved cushioned 3-point head restraint system from an ergonomics' viewpoint, but head restraints 30 also provide communications to the subject from the MR operator, relaxing music or other entertainment to the subject, and hearing protection by passive or active sound suppression means. Audio input into the head restraints 30 may be by cable, optic fiber, sound tube, or wireless means.

As can be seen from FIG. 3, head restraint earpieces 30 can be positioned in any direction to accommodate the size of the subject's head. Furthermore, head restraints 30 and head cushion 31 may come in a variety of sizes for use on a variety of subjects. Head restraints 30 and head cushion 31 would be chosen, depending on the subject's head size to ensure that the subject's head is held snugly in coil 24 to prevent motion, but not so snug as to cause pain. Further, because head restraints 30 and head cushion 31 are compact they do not crowd coil 24, thus allowing the use of a smaller more efficient coil while reducing any feeling of claustrophobia. Other methods of adjusting head restraints 30 and head cushion 31 are contemplated, such as having cushions that can expand and contract to the subject's head by simply rotating them in a clockwise-counterclockwise motion, cams, or other means without departing from the spirit of the invention. With further reference to FIG. 3, guiding slots 32 are shown. Guiding slots assist in assuring mutual alignment between top section 28 and bottom section 26.

With reference to FIGS. 4 & 5, an I/O device of the present invention is shown. I/O device 40 can be any type of I/O device including but not limited to mirrors, prisms, video monitors, LCD devices, optical motion trackers, etc. In one embodiment I/O device 40 has a front mirror 44 and a rear mirror 46 facing the front and rear of coil 24 respectively and is mounted on track 42 over the subject's face. I/O device 40 can then be adjusted to multiple positions, directions, and configurations without moving the subject. Further, in contrast to prior systems where the outside radius of the coil is increased by mounting I/O device(s) on top of or extending from the top of a coil, I/O device 40 is mounted wholly or in part within the radius or outside dimensions of coil 24. It can be seen from FIGS. 4 & 5 that I/O device 40 is particularly well suited for mounting inside open window 29 (discussed in more detail above) above the face in coil 24. I/O device 40 can be moved along track 42 from one end of the coil to the other. By sliding I/O device 40 along track 42, it can be adjusted to any subject's useful viewing angle, including looking forward or backward. For example: receiving visual information projected to the subject from the front or the back of the MR magnet (discussed in more detail below). The versatile and low profile construction of I/O device 40 allows for coil 24 to be used in close fitting head only MR systems, and in head gradient inserts used in whole body MR systems. Further, it is contemplated I/O device 40 could be replaced or complemented by similar platforms to perform other I/O functions such as positioning temperature, air, oxygen, anesthesia, IV tubes, or the like relative to a subject's mouth or nose. It is further contemplated that input/output device 40 can be any visual, olfactory, gustatory, or auditory transducers providing two way communication or stimulus. I/O devices can also be used for delivery of therapy, robotic execution of surgery, and physiological monitoring including temperature, blood pressure, respiration, EEG, EKG, etc.

With respect to FIG. 6, a front view of a resonator is shown. As discussed above, back planes on RF coils function as an RF mirror to extend the uniformity of the coil's transverse RF magnetic field along the rotational or “z” axis of the coil. The lack of end rings on a TEM coil further enhances the field extent on the z-axis. A back plane or end cap can be used in coil 24 located within back wall 62 to make the coil shorter on the z axis, and therefore more ergonomic, better shielded, and more electrically efficient coil for a desired field of view. In coil 24 for example, back wall 62 of coil 24 housing a back plane makes it possible to build a coil short enough to fully expose a subject's mouth, and make the coil more efficient at higher frequencies, while still covering the whole head field of view desired for a standard head coil. In contrast, a conventional cylindrical birdcage head coil without an end cap may be twice as long, less efficient at high frequencies, and more prone to promoting claustrophobia. A back wall in a head coil is more desirable for coil performance and ergonomics on the “mouth” end of the coil.

Visual signal projection is often performed from the rear of a magnet and through the back of a coil to mirror or prism systems mounted above the subjects' eyes. Blocking this access with a coil back plane or endcap therefore prevents visual signal projection. The present invention solves the rear magnet access problem; at least in part by providing a substantial channel 60 in back wall 62 of coil 24. Opening 60 is located high in coil 24 to minimally affect the imaging performance in the head area of coil 24 while giving maximum access for rear visual projection systems. Therefore, opening 60 allows the coil 24 to preserve the advantages of a closed end coil, while allowing for most of the benefits of an open-ended coil. Further, channel 60 provides general medical access for temperature, air, oxygen, anesthesia, IV tubes, EEG leads, physiological monitors, or the like.

The tuned TEM resonator of the present invention is exemplified by a transmission line tuned coaxial cavity resonant in a TEM mode. The coaxial line tuning elements correspond to the “slotted” hollow center conductor of this coaxial cavity.

In FIGS. 8 a and 8 b, the TEM cavity volume coil is shown in the form of a reentrant cavity 121 such as is used for klystrons and microwave triodes (8). The cavity is reentrant in that its conductive boundaries 122, 123, 124, 125 and 126 extend into or reenter the volume encompassed by the cavity. Using transmission line theory, approximations of the distributed impedance coefficients R, L, C, the fundamental TEM mode resonant frequency, and the resonant Q of this cavity are made. The coaxial cavity is similar to a coaxial line shorted at two ends and joined in the center by a ring capacitor C_(c)′ and having the dimensions o.d.=2b_(c)′ i.d.=2a_(c) length=2l. The input impedance to each low loss, shorted coaxial half cavity is given by Z _(in) =Zo tan h(α+jβ)/   (1) The characteristic impedance for this coaxial cavity is derived from Eq. (2). Z _(o) =√L/C=(η/2π)(ln b/a) for η=√(μ/ε)   (2) For a coaxial cavity whose outside radius is b_(c) and whose inside radius is a_(c)′ Z _(oc)=(η₀/2π)ln(b _(c) /a _(c))   (3) Z _(inc) =Z _(0c) tan h(α_(c) +jβ _(c))|, α_(c) ≈R _(c)/2Z _(0c)   (4) for α=0, Z_(inc)=Z_(Oc) tan β_(c)l   (5) For Z_(inc)=X_(inc) Eq. (12), the distributed inductance L_(c) of the low loss cavity is: L _(c)=2X _(inc)/ω2Z _(0c) tan h(α_(c) +jβ _(c))l/w   (6) For the low loss coaxial cavity, L _(c)=2Z _(0c) tan(β₀ l)/ω=2Z _(0c) l/u ₀   (7)

Compared to a lumped element coil circuit enclosing a given volume, the inductance Lc of the coaxial cavity containing the same volume is significantly lower. The center gap series capacitance Cc required to resonate this cavity at the design frequency f=ω/2π is: C _(c)=½ωX _(inc)=½ω(Z ₀ tan h(α_(c) +jβ _(c))l)   (8) And for the low loss approximation, C _(c)=1/(2ωZ ₀ tan β₀ l)   (9)

This center conductor gap capacitance could be supplied in lumped elements or by a capacitive ring 127 as pictured in FIGS. 8 a and 8 b. Stray capacitance Cs between the inner and outer walls of the coaxial cavity contributes a small fraction of the value Cc. Cs ultimately limits the cavity's self resonance frequency which is substantially higher than that of the lumped element coil of the same volume; a cavity of human head coil size will resonate above 500 MHz, for example. The stray capacitance for the lossless coaxial cavity is approximated by, C _(s) =πεl/ln(a/b)   (10)

The fundamental TEM mode resonant frequency f₀ of the cavity given by Eqs. (9, 10) is: f ₀=1/(2π√(L _(c) C _(c)))   (11)

The series conductor resistance R_(c) in the cavity is determined by the frequency dependent surface resistance R_(s): R _(c)=(R _(s)/2π_(c))(1/a _(c)+1/b _(c))2l, where R _(s)=√(ωμ₀/2σ)=1σδ  (12)

Shallow skin depth δ of current flux in a good conductor τ=δ(10⁷), S/m makes for the requirement of a large surface area of cavities for minimizing R. The skin depth, δ, of copper at 100 MHz, for example, is 0.0066 mm. δ=1/√(πfμmuσ)   (13)

The small, high frequency skin depth dimension however allows the use of very thin foil or surface deposited conductors which adequately conduct (and contain) RF currents and fields, but effectively attenuate low frequency eddy current propagation as induced by switching B₀ field gradient currents in the MR application. The characteristically high resonant Q_(rc) of the cavity is: Q _(rc)=βc/2αc=2πf ₀ Z ₀ /R _(c)−_(c)   (14)

Although the optimum TEM mode Q occurring for the b/a ratio of 3.6 is not readily achievable in head and body coil applications in the meter bore magnet, practical coil dimensions allow for unloaded Q values in excess of 1000. The advantageous properties of decreased inductance, decreased resistance, increased frequency, high Q, and serf shielding for the coaxial cavity should now be clear.

To permit TEM mode magnetic field propagation in the utility center of the coaxial cavity, the hollow center conductor (reentrant wall with capacitive cylinder), must be slotted (1, 2). Unshielded lumped element capacitors or capacitive plates bridging the cavity's slotted center conductor “leak” to the conservative electric (E) field largely stored within these capacitors. Problematic stray E fields, however, which adversely affect the coil's tune, match, and phase stability as well as efficiency, can be better contained by using N coaxial line elements as tubular, shielded capacitors 129 (3), as in FIG. 9 b. The conservative E field for the resulting TEM resonant cavity is thus largely contained within the dielectric regions between the floating outer conductors 130 of the coaxial elements, and the reentrant center conductors 131 which are interrupted or split at 132, but are otherwise continuous with the cavity 121. (FIG. 9 b) The coaxial tuning element used is similar to a pair of open ended coaxial lines joined in the center by a continuous outer conductor.

For the fundamental TEM mode resonance, each mirrored pair coaxial element is in balanced series resonance with the cavity. The current waveform peak amplitude is centered on these balanced elements, and effects a transverse virtual ground plane which bisects the tuned cavity. A desired transverse B₁ field maximum and an E field minimum are thereby generated within the cavity center as desired.

The TEM cavity resonator is tuned to the design frequency by adjusting the reactance (both L and C) of the line elements 9. Gross adjustment is managed by dimensional design of the elements and the cavity. Fine tuning is performed by manipulating the center conductor gaps in the elements, i.e. positioning the center conductors to appropriate insertion depths.

The transmission line element tuned coaxial cavity according to the invention is the basis for high frequency, large dimensioned volume coils for MR applications, and can be briefly characterized as a “tuned TEM resonator”.

Transmission line theory (7) provides the design equations for the TEM resonator. The input impedance to each open coaxial half element is given by Eq. (15). Z _(in) =Z ₀ cot h(α+jβ)l   (15) and its characteristic impedance is derived from Eq. (2). For the input impedance Z_(in)=X_(ine) and characteristic impedance Z₀=Z_(0e′) the distributed capacitance C_(e) for each of the coaxial tuning elements is: C _(e1/2=ω) X _(ine)=1/(2ωZ _(0e) cot h(αe+jβe)l)   (16)

The distributed capacitance of a series pair of lossless open line segments is easily calculated using jZ₀ cot ≈l for approximating Ce Ce=tan βel/2ωZ _(0e) =l/2Z _(0e) u=πε _(e) l/ln(b _(e) /a _(e))   (17)

A coaxial tuning element of the cavity length 2l, FIG. 9 b, is constructed for a desired C_(e) by choosing the appropriate dimensions for the center conductor radius a_(e) and the outer conductor radius b_(e). The dielectric material for the elements is typically not air, therefore ε_(e)=ε_(r)ε₀ where the relative permitivity for commonly used Teflon is ε_(r)=2. The distributed inductance L_(e) for each coaxial element can be similarly derived from Eq. (15) for L_(e)=2X_(ine)/ω, and approximated by: L _(e)≈(Z _(0e)2le/u)=Z _(0e)√(μ₀ε_(e))2l   (18) From Eq. (12), the resistance R_(e) per element is: R _(e)=((1/δσ)/2π)(1/a _(e)+1/b _(e))2l   (19)

The total series inductance L_(t′) capacitance C_(t′) and resistance R_(t′) for an N element tuned TEM resonator are: L_(t)≈L_(c)+L_(e)/N   (20) C_(t)≈NC_(e)   (21) R_(t)≈R_(c)+R_(e)/N   (22) Resonant frequencies are: f _(r)=ω₂/2π=βu/2π=nu/4l=n/(4l√(LC)), n=integer   (23)

In the approximations for L and C above, small amounts of mutual inductance and stray capacitance in the TEM resonator structure were not considered. By Eqs. (20,21, and 23) the TEM mode resonance for the tuned TEM resonator is: f_(0t)≈1/(2π.pi√(L_(t)C_(t)))   (24) The Q factor for the TEM resonator is: Q_(t)≈2πf₀L_(t)/R_(t)   (25)

When coupled inductively or capacitively to a matched transceiver network, the quality factor becomes Q/2 for the circuit loaded TEM resonator.

TEM resonator modes: The tuned TEM resonator is a closed-ring periodic delay line similar to a traveling-wave magnetron oscillator (9).

In the traveling wave type oscillation, the mode M dependent phase difference φM between the electrical oscillations of N successive tuning elements is such to produce a rotating AC field or traveling wave periodic with ^(T) _(M) in the interaction space between the elements and the cavity of the resonator. φ_(M)=2πM/N=β ₀ ^(T) _(M)   (26)

The traveling wave propagates in the azimuthal direction at an angular phase velocity ω_(M) for the fundamental harmonic of mode M and phase constant β₀ where angular phase velocity ω_(M) equals the resonant or eigen frequency of the corresponding mode. +ω_(M)32+β₀dφ/dt   (27)

In the pass-band of the resonator, +φ<π, therefore from Eq. (27), 0<M<N/2 for the integer M. (N/2+1) resonant modes are possible in the tuned TEM resonator. M=Nφ _(M)/2π  (28)

The fundamental modes and corresponding resonant frequencies of the eight element tuned TEM resonator are graphically described in FIG. 10. The ordinate y is the unitless “retardation” ratio of the free space propagation velocity to the “slow-wave” angular velocity of the closed delay line resonator of radius a. y=c/aω=Mλ ₀/2πa=Mλ ₀ /N _(T)   (29)

The abscissa is the ratio of the free space wavelength λ₀ to the modal period T _(M)=2πa/M for the resonator. The curves y=f(λ₀/T) for constant M/N are constant lines through the origin. The frequencies of the different fundamental modes are determined by the intersections of these constant mode lines with the dispersion curve: c/aω=f(λ₀ /T)   (30)

Because the angular phase velocity ω has positive and negative components (traveling waves propagate in two directions around the closed-ring resonator), separate dispersion curves of positive and negative phase φ may exist resulting in more possible frequencies for the tuned TEM resonator, N in total.

The lowest frequency corresponding to M=0 (the cyclotron frequency mode) is the self resonance of the tuned TEM resonator Eq. (24). For this frequency with all tuning elements oscillating in phase, φ=0°. The highest frequency and upper boundary for the fundamental modes corresponds to M=N/2, the π mode. In this mode all tuning elements are in phase opposition with adjacent elements, φ=+180°. A single frequency standing wave results.

The remaining (N/2−1) modes of resonance are degenerate doublets for imperfect TEM resonator symmetries. A slight departure from circular symmetry in the resonator will cause+dispersion curve separation resulting in degenerate mode splitting. The azimuthal current distribution as a function of φ in the resonator elements can be generalized for an imperfect coil as a Fourier series of positive phase (co-rotating) and negative phase (counter-rotating) traveling waves of unequal amplitude and phase, I=Σ ₁ ^(∞)(A _(M) ^(cos)(ωt−Mφ+δ)+B _(M) ^(cos)(ωt+Mφ+ξ))   (31) where δ and ξ are arbitrary phase constants. For perfect circular symmetry where A=B, and δ=ξ, the doublets converge to a single frequency for each respective mode. As coupling between the tuning elements decreases, the modal resonances converge toward a single frequency approximated by Eq. (24).

Mode M=1 corresponding to φ=2π/N is the TEM mode of choice for the clinical MR application. This mode produces a transverse B₁ field whose maximum magnitude and homogeneity are coincident with the central transverse virtual ground plane of the tuned TEM volume coil. The 2π/N mode can be driven in quadrature for improved MR coil transmission and reception efficiency. This M=1 mode is closest to the single cyclotron mode (M=0), and is easily identified in non optimized coils as the lowest frequency split resonance.

According to the invention, if only eight elements of the resonator are tuned for a given frequency, the other eight are tuned for a different frequency, i.e. the TEM resonator can be double tuned by tuning even and odd elements respectively to two widely different frequencies (6). Two resonance groups then result of (N/4+1) modes each. Each resonance group consists of 2 single resonances separated by (N/4+1) degenerate double resonances.

The second mode of each group generates the desired transverse B₁ field for the MR application. The double tuned TEM resonator so described is similar to the “rising-sun” magnetron oscillator (9).

These are shown in FIGS. 15 and 18. Since FIG. 18 in effect contains FIG. 15, the following description of my invention will be mainly in terms of FIG. 18.

According to my invention, the same coil structure can allow operation at two or more frequencies. For example, the FIG. 15 coil can provide fields at either of the commonly used values 70 MHz and 178 MHz. That is, while the 16 elements of FIG. 15, as a single set, can be tuned so that the coil can operate well at any single frequency in the corresponding range, e.g., (70-200)MHz, the elements can also be tuned so that the coil can operate well at either of 71 MHz and 175 MHz, or other frequency pair in that range. Thus, 8 of the 16 elements, preferably, every other one, can be adjusted to provide operation at 71 MHz, and the remaining 8 can be adjusted to provide operation 175 MHz. Such adjustments do not interact, because no element of one set is closely enough coupled to an element of the other set, that adjustment of the impedance of an element of the said one set, can significantly effect impedance in the said other set.

Of course, in providing multiple frequency operation, it is necessary to provide different values for other parameters, such as B₁. However, the coil of my invention can accommodate such different values by having corresponding sets of elements, which sets, once tuned, provide the desired frequencies without further adjustment of any elements, and without alteration of the physical configuration of the coil itself. In effect, then the coil of my invention is as many coils as there are frequencies for which the elements of my coil are tuned.

As will be seen from FIG. 18, my multiple tuned TEM resonator design, like the single frequency form of FIG. 15, uses 16 elements. However, these are divided into two groups of 8, each of which is mounted for adjustment independent of the other, by adjusting mechanism shortly to be described.

In practice, each group is tuned to some desired frequency by appropriately varying the depths of insertion of the center conductors, thereby fixing the elements' distributed impedances.

In use, one set or the other provides the desired field, and if necessary, is fine-tuned, just as if only 8 of its 16 elements are present. More generally, if there are n elements in all, then m thereof can form a set, thereby leaving (n−m) elements from which to form one or more additional sets.

Indeed, one will be able, in general, to provide k tunings, where k, the number of sets can be greater than 2.

Turning to FIG. 18, cavity 141, corresponding to cavity 121, FIG. 9 a, is essentially a plastic cylinder 142 having a circular plate 144 and an end ring 145 fixed thereto, these three elements being provided with a conductive foil on its inside, so as to provide the conductive cavity configuration indicated in FIGS. 9 a and 9 b. Ring 24 allows a body member, such as the human head, to be inserted into the cavity.

Like cavity 121, the cavity 141 is provided with transmission line elements 149, like elements 9, but being 16 in number. In order to provide more than one tunable frequency, two, say, for simplifying illustration of the present invention, a pair of circular non-conductive plastic plates 146 and 147 have the center conductors 150 of the elements 149 affixed thereto. In this case, every other conductor 30 is affixed to just one plate. Thus, plate 146 is affixed to the center conductor 30 of a set of elements 149 corresponding to frequency A, and plate 147 is affixed to the center conductors of the remaining elements 149, which correspond to frequency B. The outer conductors 151 of all 16 elements 149 are fixed to plate 144 and end ring 145, and are electrically continuous with the metal foil on cylinder 142, plate 144, and end ring 145.

The conductors 150 are fixed in position by collet clamps 152, which releasably secure the center conductors 150. Clamps 152 themselves are fixed in place, as by being embedded in the respective plates, which are shown as transparent, though they could as well be opaque.

It will be evident that during resonator assembly, the depth of insertion of conductors 150 in the segments 29 can be set by loosening the collet clamps, then individually adjusting the depths of insertion of conductors 150 until by actual measurement a resonant condition exists when RF energy of the desired frequency is used to energize the coil. This tuning is coarse, but at this point, the collet clamps are set to fix the depth of insertion of conductors 150. However, plate 147 can be translated along its axis (which is also the axis of cavity 141), in order to move all 8 conductors simultaneously, so as to vary their depth of insertion, by equal amounts.

(This may be taken as a description of the construction and operation of the single frequency resonator of FIG. 15. That is to say, in FIG. 15, the only difference is that the 16 center conductors 150 have their depths of insertion adjusted, just as in FIG. 18, 8 conductors are so adjusted, in order to tune to the desired frequency.)

The remaining 8 center conductors in FIG. 18 are fixed to the plate 147 by collets 32, at their outer conductors 151. As with their 8 fellows, their depths of insertion are adjusted also, but so as to tune the coil to a different desired frequency. As before, collet clamps 152 releasably fix the conductors 150 in a circular plate 147 again of transparent plastic. Like plate 146, plate 147 can be translated along the cavity axis, thereby to vary the depths of insertion of the corresponding 8 conductors simultaneously, and by equal amounts.

Various mechanical movements cam be used for translating the plates 146 and 147, and indeed they can be moved directly by hand since the conductors 150 can have something of a friction fit in the dielectric of the elements, and in any event, the plates can be clamped in place by obvious means, not shown.

Preferably, I provide a simple screw mechanism, which acts colinearly of the plates' axis. Due to the symmetry of the arrangement, the plates cannot cock, and screw threading inherently provides clamping.

In FIG. 15, such screw mechanism 153 is just that: a screw 154. The screw 154 has its outer end terminated by a knob 155 for turning it, and has its inner end journaled at 156 in plate 144. The journal 156 may be any suitable hardware rotatably securing the end of screw 154 in plate 144, so that when knob 155 is turned, the screw 154 will rotate but will be prevented from translating along the coil axis.

Screw 154 passes through plate 157, which corresponds to plate 146, via a threaded bore (not shown) in the plate, the bore being coaxial with the coil axis. Turning knob 155 therefore causes the plate 157 to translate along the coil axis, whereby to adjust the central conductors' position simultaneously and by equal amounts.

In FIG. 18, a somewhat more complex screw mechanism 158 is provided. Mechanism 158 has a knob 159, corresponding to knob 155, in that turning it translates plate 146, but as will be seen later differs somewhat, structurally, from screw 153, though otherwise performing the same tuning function.

Corresponding to journal 156, mechanism 158 has journal 160 rotatably securing it to plate 144. Screw mechanism 158 is also threaded to plate 147 for translating it along the cavity axis.

FIG. 19 shows screw mechanism 158 in longitudinal section. Thus, corresponding to screw 154 and journal 160 of FIG. 15, in FIG. 19, a screw 161, terminating in the knob 159 at one end is journaled in plate 144 for rotation, without translation along the axis of plate 144. As shown, screw 161 is threaded into plate 146. A sleeve screw 163, in which screw 161 freely rotates has at one end a journaled portion 44 securing it to plate 146 for rotation without translation when knob 165, which terminates the other end of sleeve screw 163, is turned. The sleeve screw 163 is threaded to plate 147, so rotation of the knob 165 therefore causes plate 147 to translate along the axis of cavity 141.

In use, one first tunes the elements 149 whose center conductors are clamped in the collets of plate 146. Then one turns the other elements whose center conductors are clamped in the collets of plate 147. Since there is negligible coupling among the elements, neither turning affects the other.

The tuning features described above contemplate that, at the other ends of the transmission line segments, the initial depth of insertion of the corresponding center conductors, established in assembling the cavity, will not be changed in subsequent use. (The ring 145 will, of course, support the other outer ends of the elements 149, like the ring 24 does.) Additional tuning effect could be had by varying the depth of center conductor insertion at the other ends of the elements 149. This could be managed by an arrangement of rings corresponding to plates 146 and 147, which would serve to bodily adjust such depth of insertion, as do the plates 146 and 147. Note that one end of the cavity needs to be open for insertion of a body or body member.

In sum, then, one set or the other provides the desired field, and if necessary, is fine-tuned just as if only 8 of its 16 elements is present. More generally, if there are n elements in all, then m thereof can form a set, thereby leaving (n−m) elements from which to form one or more additional sets.

Indeed, one will be able, in general, to provide k tunings, whereby k, the number of sets, can be greater than 2.

The same approach allows the coil to be multiply tuned, in general, i.e., to three or more resonances.

TEM resonator B₁ fields: The free space magnetic vector potential contours (flux lines) for the five modes of the eight element TEM resonator are schematized in FIGS. 11 a-11 e. The mode M=1 is the obvious choice for efficient, homogeneous magnetic coupling to a central region of interest. Such free space AC fields are often approximated by the DC field Biot-Savart law. At radio frequencies beginning at about 100 MHz however, static field approximations of RF fields in human anatomy are no longer accurate. Similarly, simple homogeneous, isotropic geometries (spheres and cylinders) are not appropriate for modeling the human load.

Viewing the human body as a heterogeneous, lossy dielectric of tissue wavelength proportions, the electromagnetic propagation boundary effects of refraction, reflection and attenuation must be considered. Substantial axial eddy current shielding and orthogonal displacement current extension of the B₁ field are observed in human tissues at high frequencies. Fully time-dependent equations and complex numerical models are required for describing the high frequency coil B₁ field distribution in anatomic regions of interest. A time-harmonic magnetic field B₁/μ in a lossy, anisotropic, inhomogeneous coil-tissue system can be described by the differential form of the Maxwell-Ampere Law (10): ∇XB ₁ /μ=J _(c) +δD/δt   (32)

By Ohm's Law the current density J_(c)=σE, and by Euler's Law the electric field displacement δD/δt=δεE/δt=jωεE so that Eq. (32) can be rewritten as: ∇XB ₁/μ=(σ+jωε)E   (33)

The complex value of E can be written in terms of the magnetic vector potential A, and the electric scalar potential Ψ, such that: ∇XB ₁/μ=(σ+jωε.)(−jωA−∇ψ)   (34)

Influencing the B₁ distribution and loss in human tissues adjacent to the coil are the B₁ field induced eddy current density, J_(e)=−jωσA, and the accompanying electric field displacement current density, J_(d)=−jωεE=ω²εA for tissue specific values of σ and ε. The magnetic vector potential lines A, and the contours B₁=∇XA generated in a human head model by specified resonator element currents can be determined by solving numerically for A and Ψ in the equation: ∇X1/μ∇XA=(σ+jωε)(−jωA−∇ψ)   (35)

In FIG. 12, the Finite Element Method (FEM) is used to model a human head loaded 16 element TEM resonator operating at 175 MHz. The magnetic vector equi-potential lines A/m, for mode M=1 of the TEM resonator were numerically solved by Eq. (35). The two layers of the head were traced from a 4.1 T MR image, and represent brain and scalp/fat/skull respectively. Table values for frequency dependent σ, ε, and μ of human brain and skull/fat were assigned to the appropriate tissue layers of the model. The cross sectional view corresponding to the central transverse plane of the volume coil, is the Cartesian xy plane for the model with z being infinite. The coils 16 RF current elements are contained within a cavity's usual grounded conductive cylinder. With equal RF current amplitude in the elements separated by phase φ=2π/N, a transverse electromagnetic (TEM) field is generated within the transmission line model as shown. Note the flux line rotations present in the high frequency coil-head model of FIG. 12, but not seen in the free space/static field representation of M=1 in FIG. 11.

Calculated B₁ contours, T/m for phantom and head loaded TEM resonator models are shown in FIGS. 13 a and 13 b. Central to the current elements in FIG. 13 a, is a 20 cm human head phantom identified by the contour pattern of five concentric circles. The phantom was assigned σ, ε, and μ values of human brain. All space not occupied by the coil cylinder, elements or subject's head is free. With a 175 MHz, 2 ampere current assigned to the elements, a 10 μT B₁ field is generated in free space at the surface of the head phantom. At 175 MHz the head becomes a lossy dielectric resonator with a B₁ field distribution substantially different than that of free space. The model predicts an attenuation of the B₁ field by 3 μT (30%) in the outside ⅓ radius of the phantom. This is the expected result of eddy current shielding. The model also predicts more than a 1 μT (10%) B₁ field enhancement in the inside 1/10 radius of the head. This displacement current induced B₁ enhancement compensates for the increased shielding expected for higher frequencies such that B₁ homogeneity is adequate for imaging the human head and body in fields of 4 T and higher. FIG. 13 b presents the FIG. 12 scale model of a head within a coil which is excited with current levels required for gradient echo imaging at 175 MHz. The model predicts B₁ contours of highest magnitude to be in the frontal and occipital regions of the head due to their close proximity to the coil elements. The more distant temporal regions are lower in B₁ magnitude. The center of the brain shows the displacement current B₁ enhancement characteristic of the fortuitous coincidence of tissue σ/ε and human head electrical dimensions at higher frequencies. Also beneficial is the eddy current retarding effect of the heterogeneity of human tissue and anatomical structure. The more heterogeneous two layer model in FIG. 8 b predicts a B₁ inhomogeneity of less than +10% magnitude variation over the head compared to +15% variation over the single layer isotropic model of FIG. 8 a. Empirical observations support the predictions from the coil-head, and coil-phantom models above (2, 4, 5, 13, 14).

Alternative TEM resonator models: So far, transmission line theory was used to describe the tuned TEM resonator as a transmission line tuned coaxial cavity resonator. Alternatively, the TEM resonator can be approximated as a balanced comb-line, band-pass filter using the lumped element circuit of FIG. 14 a. The lumped elements in this circuit approximate the distributed element coefficients of the transmission line circuit. Analysis of this lumped element filter circuit model adhering to methods in the literature for “bird-cage” resonators gives inaccurate results (15, 16). My invention's more accurate approach considers the lumped element filter's distributed stripline analogue in FIG. 14 b. This network is a quarter wave (as in FIGS. 7 a and 7 c) comb-line filter interfaced with its mirrored image at the virtual ground plane of symmetry indicated by the dotted line. Each coaxial element, due to its split central conductor, therefore is a resonant half wave line (mirrored quarter wave pair, as in FIGS. 7 b and 7 c wave pair) whose bisected center conductor 11 is grounded at both ends to a cavity. The elements 9 are coupled via the TEM slow wave propagation h the cavity. The performance characteristics of this distributed structure are calculated from TEM assumptions (17).

Methods and Materials

TEM resonator construction: Single and double tuned TEM resonators have been built for clinical MR applications from 70 to 175 MHz. Prototypes have been bench tested to 500 MHz. Thus, FIG. 15 shows a 175 MHz (4.1 T) head coil. Here the tuned TEM human head sized resonator measures 34 cm o.d. (cavity) by 27 cm i.d. (elements) by 22 cm in length. The i.d. and length were determined by head size while the o.d. was chosen for compactness with some sacrifice of the optimal coil Q predicted for a larger cavity Eq. (14). The cavity itself is constructed of 1 mil copper foil 13 fitted to the inside and outside surfaces of an acrylic cylinder Eq. (13). Acrylic end members support the reentrant tuning elements and the copper foil making their continuity with the cavity. The cavity could be extended with foil on plate 144.

N.B. A “transmission line element” need be no more than a pair, or more, of conductors side by side, and AC coupled to each other by a dielectric therebetween. It is evident, therefore, that “coaxial cable” is not the only form the “elements” or “segments” may take in the process of my invention.

The tuning elements are 21 cm coaxial line segments 9 whose outer member 31 is a copper conductor whose i.d. is 12.7 mm (0.5″), and whose center conductor 30 is a bisected 6.5 mm (0.25″) o.d. copper rod. Teflon sleeve inserts (not shown) provide the dielectric between conductors 150 and 31, and are machined to serve as both a dielectric and bearing surface between the two conductors. The Teflon sleeve thickness (b_(e)−a_(e)) should be greater than 3 mm to preclude the possibility of dielectric breakdown and consequential arcing during high peak power transmitting. 5 mm Teflon spacers 15 at each end of the coax segment maintain electrical isolation between the outer conductor 11 of the element 9 and the cavity foil 13 to which the center conductor is attached. See FIGS. 7 and 8 of Roschman (3) for an exemplary element construction of this sort.

The element component diameters and the number of the tuning elements used are determined for a desired frequency and coil size by starting with Eq. (25) and working backwards solving for N, a_(e), and b_(e). Assuming the lossless case for the lines and the cavity simplifies the calculations required. Using 4N tuning elements in the design facilitates quadrature drive. Typical values for N are 12 to 16 in a human head coil and 24 to 32 in a human body coil. Homogeneity is proportional to N whereas frequency is inversely proportional.

The divided center conductors of the tuning elements are conductively connected to the cavity 121 on one end thereof by the collet clamps 152, and on the other end by copper beryllium spring gaskets, copper straps, or the like. The collet clamps allow for fixed adjustment of the insertion depths of the center conductor halves during coil fabrication. The gaskets allow for variable adjustment during coil operation. By varying the insertion depth of their center conductors, the coaxial line elements are tuned to a desired coincidence of mode and frequency.

As previously described, the center conductors on one end of the cavity are mechanically linked by a mobile plate and screw mechanism such that by turning a knob or knobs all can be adjusted in concert to tune the resonator without effecting its field symmetry. Two line elements 9 separated by a 90° azimuth angle are connected to a pair of 90° phased ports 21 of a strip line quadrature hybrid for quadrature drive of the TEM resonator. See FIG. 16 which shows one of two driven line elements for a quadrature excited resonator.

The hybrid ports are properly phased and impedance matched to the coil and its human head or body load via the reactance of variable reactors comprising variable series capacitance and/or balun circuits, not shown in FIG. 15, which, however, does show knobs 166 for varying said reactance. FIG. 18 requires an additional circuit of this sort, so knobs 167 would provide for varying reactance. The quadrature hybrids for frequencies A and B are identified by reference numerals 168 and 169. Reference numeral 170 identifies FIG. 15's quadrature hybrid.

TEM resonator optimization: Frequency tuning, impedance matching, quadrature phase isolation, B₁ homogeneity and sensitivity, and Q are among the more important performance characteristics to be optimized for any quadrature volume coil. After the TEM resonator is constructed, the first step toward optimization is to adjust all elements (2N half elements) to the equal capacitance values which tone the resonator's M=1 mode resonance to the design frequency. An RCL meter is used for element capacitance measurements. A network analyzer frequency swept reflection measurement is used to produce the return loss plot identifying the 16 element head coil's 9 resonant modes in FIG. 17. Mode 1, located at 174.575 MHz will initially appear as a double resonance as mode 2 for the non optimized coil. By an iterative method of free tuning the capacitances of individual elements (not unlike the tuning of a bicycle wheel through spoke adjustment), the mode 1 doublet will collapse into the well matched, high Q, single frequency point as shown. For the quadrature coil, the plot of FIG. 17 must be reproduced for mode 1 at each of the two drive points independently. Additionally, a transmission test should confirm better than 40 dB isolation between the quadrature drive points, at the design frequency. Maximum B₁ field amplitude should be verified on the axes orthogonal to the bisecting longitudinal planes of the coil containing the driven elements. B₁ transmission field magnitude and homogeneity are measured on the quadrature x and y axes with a directional magnetic field probe receiver. After the alignment of quadrature, well matched and isolated, high B₁ amplitude resonances at the mode 1 design frequency in the unloaded coil, the optimization process is repeated for the phantom loaded coil. The phantom electrically mimics a human head in volume and conductivity. The resonator is then fine tuned on human subjects. A stripline quadrature hybrid is finally connected to the two capacitively matched, quadrature drive points of the resonator. In the optimized coil, two superposed quadrature B₁ fields corresponding to the mode 1 frequency are measured, with peak amplitudes of 3 dB less gain than the previously measured single drive point linear fields. With all adjustments complete, the sliding center conductors of the coax segments are clamped into position at both the fixed ring and mobile plate ends of the coil. In the magnet, the resonator is tuned to different loads by turning the central knob 155 shown in FIG. 15, 46 are adjusted for precise impedance matching and 90° phase isolation between the two coil ports of the quadrature hybrid. Tune, match, and phase adjustments can readily be performed on each study.

Results

Single and double tuned TEM resonators perform efficiently from 70 to 175 MHz in human head and body applications. The Q ratio of a 175 MHz tuned TEM head coil design is a high 840/90 typical of resonant cavities. The tuning range for this tuned cavity design is arbitrarily large to an octave or better. This range facilitates the use of a given coil at different field strengths and for different nuclei. For a whole human head, 90° optimization is typically achieved with a 1 kW, 250 μsec square pulse. For each MR study performed, the TEM resonator is tuned to frequency, matched to a VSWR of 1.0 at both coil drive points, and quadrature phase isolated to greater than 50 dB, all without adversely influencing B₁ field symmetry. This In Situ optimization requires three external adjustments and less than three minutes time.

B₁ field patterns observed in phantom and human loads are consistent with the model predictions of FIG. 13. Equal element currents correlate to maximum homogeneity of B₁ field distribution in axis symmetric phantoms coaxially located within the coil. Head images from resonators with equal element currents do not show the best achievable homogeneity. The B₁ contour pattern calculated for equal currents in FIG. 13 predicts the inhomogenities in the head image of FIG. 18. B₁ coupling of the highest magnitude is in the occipital region of the head due to the head's close proximity to the coil elements. The intensity of B₁ coupling to the frontal region of the brain which is spaced further from the coil elements to allow for the nose, is less. The more distant temporal regions show the least signal intensity and corresponding B₁ field strength. The center of the brain shows the displacement current B₁ enhancement predicted. At high frequencies, a more homogeneous B₁ distribution in the head or other loads lacking perfect axial symmetry and position can be achieved by asymmetrically adjusting individual element currents while otherwise maintaining optimized performance characteristics for mode 1 of the coil. Element currents affecting higher homogeneity for a design and application can be calculated as before by numerically solving Maxwell's equations for finite-element scale models of the loaded coil. Homogeneity in the human head of 10% variation over a 15 cm d.s.v. has been achieved in practice, using a T1 weighted gradient echo sequence wherein TR=2500 ms, TE=17.5 ms, and TIR=1000 ms for a 3 mm, 512² resolution single acquisition image. Only a relatively low level 400 W peak RF prefocussed pulse excitation wave form was required for head images. This is in contrast to the exceedingly high levels formerly predicted in the literature for high field clinical imaging. High resolution definition of the transcranial vascularity is thought to be enhanced by the high field susceptibility gradient imparted by the relative paramagnetism of deoxygenated hemoglobin in venous blood. 3 mm and 5 mm slice thickness brain images of 512² and 1024² resolution showing submillimeter detail of brain vasculature and neuroanatomy have been obtained (4, 18). Excellent quality human head and body images have been shown (19).

Using the tuned TEM resonator at 4.1 Tesla, the potential for scientific studies and clinical diagnostics from anatomic, spectroscopic, and functional imaging of the brain has been convincingly demonstrated. With 400 μM in plane resolution from 3 mm slices, clinically important structures such as the basal ganglia, red nuclei, thalami and the substantial nigra were clearly visualized in 20 volunteers, potentiating image based diagnoses of neurodegenerative disorders such as Parkinson's disease (20). In 8 healthy volunteers and 7 patients with temporal lobe epilepsy, the internal anatomy of the hippocampal formation was well defined. The alveus and fimbria were resolved from adjacent cellular layers; the stratum radiatum and lacunosum were resolved from the cornu ammonis. Atrophy, normal layer disruptions, and/or T1 and T2* deviations clearly indicated the affected hippocampus in all seven patients studied (21). High resolution spectroscopic images (0.5 cc voxels) from 10 healthy volunteers and 3 multiple sclerosis (MS) patients indicates the potential for using the spatial variability of NAA, creatine, choline, and lactate across MS plaques for the diagnosis and understanding of the disease (22). In high resolution NAA images of the whole brain, the loss of NAA from small stroke penumbra is dramatic (23). The high spatial and temporal resolution detection and quantification of the amino acids glutamate and glutamine are important for mechanistic studies and diagnoses of metabolic disorders such as hepatic encephalopathy (24). High resolution spectroscopic imaging studies of 10 human subjects have been used to quantify gray and white matter metabolites in the whole brain In-Vivo (25). The tuned TEM resonator has proven effective for the application of homogeneous, high resolution 3-D cerebral activation mapping (functional imaging) of the human brain at 175 MHz (26). The preceding results and those from studies in progress, demonstrate the effectiveness of the tuned TEM resonator design for high field clinical applications.

Human in, ages and spectra obtained with an experimental 4.1 T MR system indicate the advantages gained by performing clinical studies at higher B₀ fields. These advantages of S/N, spatial resolution, temporal resolution, chemical shift resolution and the magnetic susceptibility enhancement of brain and other organ functions point to higher B₀ fields in clinical MR.

My new RF coil achieves these advantages, so it can replace coils of the present lumped element technologies which perform poorly for clinical sized volumes at higher frequencies. The distributed technology presented herein, making use of transmission lines and resonant cavities, perform well over the tested bandwidth of 70-175 MHz for human head and body coil applications. Beyond this, bench tested prototype single and double tuned large volume coils forecast successful use of the tuned TEM resonator at frequencies to 500 MHz, for human volumes, and even higher for smaller volumes.

References

-   1. H. J. Schneider, and P. Dullenkopf, Rev. Sci. Instrum. 48, 68     [1977]. -   2. H. Barfuss, H. Fischer, D. Hentschel, R. Ladebeck, A. Oppelt, R.     Wittig, W. Duerr, and R. Oppelt, MR Biomed. 3, 31 [1990]. -   3. P. K. Roschmann, U.S. Pat. No. 4,746,866 [1988] -   4. J. T. Vaughan, J. O. Otu, H. P. Hetherington, P. Noa, G. M.     Pohost, in “Book of Abstracts, Society of Magnetic Resonance in     Medicine, 11th Annual Meeting, Berlin, 1992,” p. 279. -   5. J. T. Vaughan, H. P. Hetherington, J. G. Harrison, J. O.     Otu, J. W. Pan, P. J. Noa, G. M. Pohost, Phys. Med. [1993] -   6. J. T. Vaughan, H. P. Hetherington, J. W. Pan, P. J. Noa, G. M.     Pohost, in “Book of Abstracts, Society of Magnetic Resonance in     Medicine, 12th Annual Meeting, New York, 1993,” -   7. R. A. Chipman, “Theory and Problems of Transmission Lines”,     McGraw-Hill, New York, 1968. -   8. S. Y. Liao, “Microwave Devices and Circuits”, Prentice-Hall,     Englewood Cliffs, N.J., 1985. -   9. R. Chatterjee, “Elements of Microwave Engineering,” Ellis     Horwood, Chichester, England, 1986. -   10. R. F. Harrington, “Time-Harmonic Electromagnetic Fields,”     McGraw-Hill, New York, 1961. -   11. Maxwell® Engineering Software System, Ansoft Corporation,     Pittsburgh, 1992. -   12. F. A. Duck, “Physical Properties of Tissue”, Academic Press,     London, 1990. -   13. H. Bomsdorf, T. Heizel, D. Kunz, P. Roschmann, O. Tschendel,     and J. Wieland, MR Biomed. 1, 151 [1988]. -   14. J. T. Vaughan, J. Harrison, B. L. W. Chapman, J. W. Pan, H. P.     Hetherington, J. Vermeulen, W. T. Evanochko, G. M. Pohost, in “Book     of Abstracts, Society of Magnetic Resonance in Medicine, 10th Annual     Meeting, San Francisco, 1992,” p. 1114. -   15. J. Tropp, J. Magn. Res. 82, 51 [1989]. -   16. R. Pascone, T. Vullo, J. Farrelly, P. T. Cahill, Magn. Reson.     Imag. 10, 401 [1992]. -   17. G. L. Matthaei, L. Young, E. M. T. Jones, “Microwave Filters,     Impedance Matching Networks, and Coupling Structures,” McGraw-Hill,     New York, 1964. -   18. H. P. Hetherington, J. T. Vaughan, J. W. Pan, P. J. Noa, D. B.     Twieg, R. K. Kuzniecky, G. M. Pohost, J.Magn. Reson. Imag. 3(P), 313     [1993]. -   19. J. T. Vaughan, J. Harrison, H. P. Hetherington, G. M. Pohost,     J.Magn. Reson. Imag. 3(P), 314 [1993]. -   20. J. W. Pan, H. P. Hetherington, J. T. Vaughan, and G. M. Pohost,     in “Book of Abstracts, Society of Magnetic Resonance in Medicine,     12th Annual Meeting, New York, 1993” -   21. R. Kuzniecky, H. Hetherington, J. W. Pan, and G. M. Pohost, in     “Book of Abstracts, Society of Magnetic Resonance in Medicine, 12th     Annual Meeting, New York, 1993” -   22. J. W. Pan, H. P. Hetherington, G. F. Mason, J. N. Whitaker,     and G. M. Pohost, in “Book of Abstracts, Society of Magnetic     Resonance in Medicine, 12th Annual Meeting, New York, 1993” -   23. H. P. Hetherington, J. W. Pan, G. F. Mason, S. L. Ponder, D. B.     Twieg, J. T. Vaughan, and G. M. Pohost, in “Book of Abstracts,     Society of Magnetic Resonance in Medicine, 12th Annual Meeting, New     York, 1993” -   24. G. F. Mason, J. W. Pan, H. P. Hetherington, S. Ponder, D. Twieg,     and G. Pohost, in “Book of Abstracts, Society of Magnetic Resonance     in Medicine, 12th Annual Meeting, New York, 1993” -   25. H. P. Hetherington, J. W. Pan, G. F. Mason, S. L. Ponder, D. B.     Twieg, J. T. Vaughan, and G. M. Pohost, in “Book of Abstracts,     Society of Magnetic Resonance in Medicine, 12th Annual Meeting, New     York, 1993” -   26. D. B. Twieg, J. W. van der Veen, R. K. Justice, J. den     Hollander, H. P. Hetherington, J. T. Vaughan, G. Deutsch, and G. M.     Pohost in “Book of Abstracts, Society of Magnetic Resonance in     Medicine, 12th Annual Meeting, New York, 1993” -   27. P. K. Roschmann et al., U.S. Pat. No. 4,712,067 (1987). -   28. Kemmer et al, U.S. Pat. No. 4,737,718. 1988. -   29. Mens et al, U.S. Pat. No. 4,952,878, 1990.

It will be appreciated that the present invention can take many forms and embodiments. The true essence and spirit of this invention are defined in the appended claims, and it is not intended that the embodiment of the invention presented herein should limit the scope thereof. 

1. A magnetic resonance apparatus, comprising: a coil having at least two separable sections; an input/output device; said input/output device located within an open face area in said coil.
 2. The apparatus of claim 1, wherein said input/output device is selected from the group consisting of visual transducers, olfactory transducers, gustatory transducers, or auditory transducers to provide two way communication.
 3. The apparatus of claim 1, wherein said input/output device is mounted generally above a subject's face.
 4. The apparatus of claim 1, wherein said input/output device provides positioning for temperature, air, oxygen, anesthesia, and IV tubes to a subject.
 5. A TEM coil, comprising: an input/output device; said input/output device located within an open face area in said coil.
 6. The TEM coil of claim 5, wherein said input/output device is selected from the group consisting of visual transducers, olfactory transducers, gustatory transducers, or auditory transducers to provide two way communication or stimulus.
 7. The TEM coil of claim 5, wherein said input/output device is mounted generally above a subject's face.
 8. The TEM coil of claim 5, wherein said input/output device provides positioning of temperature, air, oxygen, anesthesia, and IV tubes to a subject. 